Crossarm insulator pin auxiliary mounted passive all fiber electro-optical current sensor

ABSTRACT

A device for installing an all fiber optoelectrical transducer on the base of a pin insulator column, such that the device mounts to the insulator pin column in a bushing style of concentric attachment and enables retrofits of said device to existing transmission &amp; distribution bushing insulator equipment. A rigid and solid mechanical support region contains a hollow bushing attachment point at a center location, and radiates outward and bonds solidly and statically to a hollow toroidal conduit, which houses optical wave guides, terminating at auxiliary connection ports, located on the exterior of the hollow toroidal conduit region, while hollow conduit support arms extend from the exterior conduit ring to a power conductor region, and integrate with optical connection ports located on static support stands, where the optical ports interface with a detachable and flexible fiber loop transducer, which surrounds an energized power conductor.

BACKGROUND OF THE INVENTION

Energized high voltage power lines and fiber optic waveguides have proven to function in close proximity without interference, and this relationship is exploited in applications such as optical power ground wire (OPGW), where high-speed fiber optic conductors are embedded within overhead electric transmission wires and routed along the same conductor path.

For electrical power system supervisory control and data acquisition (SCADA), visibility and monitoring resolution are dependent on sensor distribution and range. Along high voltage distribution lines, increasing the resolution of line current monitoring can yield advantages.

Fiber optic current sensors measure using optical materials with a non-zero Verdet constant with Faraday phase rotation, which describes the rotation of polarized light waves in the presence of an electromagnetic field, with the degree of rotation proportional to the magnitude of the proximate field:

θ[rad(T*m)]=VBL   Eq.1

Where V is the Verdet constant of the optical sensing material, B is the Magnetic Field Strength, and L is the path length of the optical sensing material.

To measure current in a linear conductor with a common mode differential element, fiber current transducers (CTs) transmit counter-propagating polarized light waves around the electrical conductor in a loop, and then calculate the relative polarization angle phase displacement or shift between the two counter-propagating waves after traversing a path around the energized electrical conductor. This common mode differential measuring scheme is robust to noise and signal interference resulting from vibration or stray EMI, as these common mode effects are cancelled at the measuring output through subtraction. By measuring the initial phase rotation of the two counter-propagating polarized light waves and then measuring their relative phase displacement after being guided around an electromagnetic field, the strength of the field can be calculated using algorithm-based microprocessor instruments. The governing equation which relates conductor current to the phase displacement induced in a polarized light wave is described as:

Δθ=(VNI)   Eq. 2

Where V is the Verdet constant, in units of radians per ampere, N is the number of fiber turns in the transducer loop, and I is the current, in unites of Amperes. The Verdet constant is wavelength-dependent, and for a wavelength division multiplexing scheme the calculations of electrical current from the phase displacement or change in rotation angle of polarized light waves would be adjusted based on the Verdet constant for the wavelength used for a specific sensor. For a SCADA microprocessor capable of receiving polarization phase angle displacement data from the polarized light waves, the current is calculated as:

$\begin{matrix} {I = \frac{\Delta\theta}{VN}} & {{Eq}.\mspace{14mu} 3} \end{matrix}$

From the prior art, it is clear that all-fiber current transducers have been perfected with high-accuracy while experiencing no saturation limitations and having much lower mass than iron-core electromagnetic current transducers, which rely on a finite number of magnetic domains within the atomic structure of a ferrite core to store primary current information in the format of magnetic flux, with hysteresis due to a 60 Hz cycling of magnetic polarity, with an integration of this process as mapped on the B-H curve yielding a non-trivial energy loss for such electromagnetic current transducing devices. Conventional electromagnetic iron-core current transformers have accuracy limitations based on finite flux storage capacity, and past the “knee” region of an accuracy curve experience saturation, where the reproduced secondary current from the CT current does not accurately reflect the primary sensed current. All fiber optical current transducers do not experience these disadvantageous performance limitations, and have a theoretically unlimited bandwidth for current sensing, which is a strong motivation for their adoption into power systems for SCADA purposes.

High voltage distribution lines in many areas do not have significant SCADA visibility, although line-clamped wireless induction-based current sensors are a recent development. Such sensors are limited in range by RF communication constraints, such that it is not clear how they could be effectively deployed in mountainous and forested areas, where line of sight wireless signal transmission limitations are common. The galvanic connection between the sensor and the power line for induction current-sensing and static mass support purposes also raises question of performance in high-fault duty scenarios, where the sensor electronics may themselves be destroyed by a high-fault current, rendering their SCADA capabilities useless.

It is therefore desirable to design a method for installing all-fiber optical current transducers onto high-voltage distribution power lines, such that distribution substation line control relays could access real-time, high-resolution current data for the entire line. Time domain reflectometry is commonly used for fault location sensing on transmission lines, as the faulted-zone impedance change causes a reflection boundary which enables simple time-of-flight calculations to determine the exact fault location. On a distribution line, it would be desirable to know the continuous current distribution at all line sections under normal, non-faulted conditions, with the ability to reproduce fault currents at specific locations when they occur. A line to line or line to ground fault on a distribution line will automatically open an upstream interruption device, which precludes time-domain fault locating due to the open circuit. With high resolution real time current sensing, the first few wave-cycles of a given fault current could be relayed to a SCADA monitoring station via the line substation's line monitoring relays, with an exact geographic fault location. From the existing art on the subject of all-fiber optical current transducers for power system applications, it is not clear how such devices could be feasibly deployed on high voltage distribution power line circuits, given the design constraints, which include the continuous cable conductors which should not be broken or spliced, environmental exposure to wind and water, the sparsity of mounting locations on a primary cross-arm, and the electrical code prohibition against the presence of secondary-voltage conductors on a primary voltage cross arm. It is therefore the purpose of the present invention to enable the deployment of all-fiber optical current transducers on distribution lines, subject to the physical design constraints inherent to distribution circuits.

SUMMARY OF THE INVENTION

The present invention provides a contained and complete solution for mounting a fiber optic loop current sensor on a distribution power line at the primary voltage level, by attaching to the base of the insulator support column mounted to the crossarm.

The fiber loop has long rigidly reinforced ends, to prevent stress of the fiber at the connectorization points. These rest on a support base and plug in to recessed weatherproof plugs. This enables the fiber transducer to be installed around an existing conductor. The fiber loop is contained within a waterproofed and flexibly armored jacket. These features prevent mechanical and environmental stress on the fiber loop. Because the electromagnetic field under measure varies at a rate of

$\frac{1}{r^{2}}$

with distance, where r is the radius extending in any polar orientation orthogonal to the conductor surface, it is necessary that the transducer loop be centered around the conductor, such that the polarized light waves traversing the loop path maintain a constant distance r from the conductor center. For this reason, the optical connection ports and their associated support stands, where the reinforced ends of the fiber transducer plug in to create a closed loop path around the conductor, are located at a height below the conductor such that their vertical displacement from the conductor center equals the radius of the transducer loop. If the support stands and associated optical ports are then horizontally oriented such that the conductor is equidistant between, then the conductor is centered within the transducer loop and the aforementioned condition for accurate Faraday rotation is satisfied.

The sensor stand contains internal fiber optic routing which connects the power line mounted fiber sensor loop to the base of the insulator support column, where transmit and receive ports link with auxiliary signal sources and sinks. The present invention features a center mounting location for bushing-style attachment to an insulator pin, and is designed to rest on a flanged surface of an insulator pin which has been fabricated with a flanged support base for the stand, on top of which the insulator columns are then stacked. This feature exploits the mechanical strength of this location and also allows for efficient installation of the sensor during planned insulator and cross-arm replacements, which occur regularly on power utility maintenance schedules.

Pole mounted sensors connect passively to the main horizontal data link, which connects all sensor locations, with a bi-directional optical coupler, located within a pole-mounted patch panel. Bend-insensitive fiber can be routed vertically, through conduit, to the primary conductor crossarm, to plug in to a sensor at the base of the insulator support column.

An advantage of the device is that it requires no active power to operate, as all signal power is provided from the central SCADA laser transmitter via the high-speed horizontal backbone using the passive optical signal network architecture.

To implement wavelength addressing for sensor identification, optical wavelength channel filters are placed in series with the bi-directional optical coupler vertical fiber riser branches, and are tuned to the specific wavelength in the channel indexing spectrum which has been assigned to a particular sensor, such that each sensor only passes one wavelength channel band from the transmitted wavelength spectrum of the horizontal datalink through its loop, and through the assignment of unique wavelength channels to different sensors, the received polarized spectrum data which is transmitted back to the SCADA photodetector receiver can be attributed to individual sensor locations, based on dense wavelength division multiplexing of the transmitted signal from the SCADA receiver along the horizontal data-link.

Power lines feature inductive reactance due to a non-zero value of L Henries resulting from their electromagnetic physical parameters. When considering the power line as a charged inductor, with energy stored in a surrounding magnetic field proportional to flux density, under electrically energized conditions the voltage can be modeled as a first order inductive element, where

${V_{L} = {L\frac{{dI}_{L}}{dt}}}.$

For fault conditions, such as in line-line or line-ground, different impedance networks exist which will alter the fault current value depending on the fault source voltage, but the inductor current time derivative term is excited by large fault current, as this represents a high and fast departure from steady state line current conditions, which induces a transient voltage, with time constant depending on the inductance magnitude and the resistive damping of the faulted line circuit. This imposes a DC offset on the line current during the initial sub-transient reactance period of a fault, lasting only a few cycles. Supposing the persistence of DC offset conditions for 3 cycles of 60 HZ fundamental, a Faraday rotation magneto-optical transducing network pulsing at mega- or giga-bit transmission rates has a relative eternity of time in which to detect the DC offset at the earliest stages of a fault. While calibrating optical current transducers for protection-class and metering-class accuracy is a serious consideration in many conventional optical CT applications, for immediate fault sensing on distribution voltage power lines, an exaggerated error rate of even 20% in the DC-offset measurement for fault current would be irrelevant to the success outcome of the binary detection task of fault location sensing in distribution or transmission power line networks.

Linear polarized light exists in two orthogonally split and transversely opposed modes, travelling along longitudinal and latitudinal axes within a waveguide medium. Birefringence describes the difference in refractive index for the perpendicular axes which the linearly polarized and split light modes travel along. Because the two axes which the linearly polarized light modes travel along have different indices of refraction, one of the linearly polarized light modes will travel faster than the other, such that a “fast” and “slow” axis is said to exist. Because the linearly polarized light modes travel at different speeds, they arrive at a destination at different times. To account for this difference in arrival time between the two polarized light modes, a differential group delay element, hereafter referred to as DGD, describes the time or distance separation between the two linearly polarized modes, as observed from an arbitrary measurement location.

If we consider the “fast” and “slow” orthogonally opposed axes of polarized light mode travel as the bounds of variation of index of refraction within the optical waveguide medium, then intuition tells us that, as a linearly polarized light mode rotates its path trajectory toward the “fast” axis, it will speed up, and as a linearly polarized light mode rotates toward the “slow” axis, it will experience a decrease in velocity.

The influence of a surrounding electromagnetic field, acting on a linearly polarized light mode travelling within a waveguide optical medium with a non-zero Verdet constant, will cause rotation of the light modes about the orthogonal polarization axes previously described. To observe the magnitude of rotation, we need only measure the change in relative velocity between the two modes, as expressed by a change in their differential group delay element, or delta Tau (Δτ). Polarization dispersion meters can measure this differential group delay element for purposes of fiber medium characterization, and an algorithmic conversion formula can convert the differential group delay element measurement to an inference of polarization angle change, which is directly applicable to the calculation of current magnitude corresponding to the flux density of the electromagnetic field which induced the linearly polarized light rotation.

In one embodiment of the present invention, linearly polarized light, easily generated through simple mechanical means, could be transmitted across a polarization-maintaining fiber medium, with a measured and known orthogonal degree of linear polarization, such that for a given sensor location, at a certain distance from the transmitting location, a predicted and expected differential group delay element is said to exist between the two linear polarized light modes, proportional to the difference in index of refraction between the two axes within the fiber optic medium, and the distance to the sensor location.

When said linearly polarized light modes reach the sensor loop, they enter a fiber medium which is not polarization maintaining and travel a complete path around an electromagnetic field of significant flux density. It is expected that both linear modes will experience a similar degree of rotation, and that this will exert opposite effects on the velocity of each, such that the previously faster mode will slow down, and the previously slower mode will speed up, as the modes which were previously orthogonally polarized at the extreme bounds of fast and slow IOR axes rotate away from the perpendicular axis positions which these extreme IOR bounds represent. Assuming that the variation of IOR between the two fast and slow orthogonal polarization axes is fully mapped and can be expressed as a continuous function, or piece-wise continuous when accounting for asymptotic singularities which could exist within the medium, then translating a change in differential group delay element, as measured for a returned linearly polarized pulse from a forward sensor location, to a degree of relative polarization angle rotation between the two modes, is possible, and is the theoretical basis for the functional purpose and operation of the present mechanical invention.

To measure the change in relative polarization angle between two linearly polarized light modes, resulting from their traversal around the electromagnetic field of an energized conductor, known waveguide birefringence can map the measured differential group delay element of the received linearly polarized modes to their relative polarization angle rotation. All fiber links within the network are polarization maintaining, except for the transducer loop, which theoretically ensures noise immunity, such that all changes in polarization angle for light pulses are due to the Faraday rotation effect based on the conductor's electromagnetic field. Where birefringence describes variable indices of refraction for light modes at different polarization angles within the fiber transmission medium, the differential group delay element between the pulses, over a known linear distance, can be used to calculate the indices of refraction seen by the polarized light modes, to account for their relative linear displacement. If the polarization-angle dependent birefringence is mapped as a continuously variable function for all polarization angles, then the change in differential group delay element measured between the transmitted and received linearly polarized light modes can be used to directly infer the change in relative polarization angles, which rotated the light modes onto optical path trajectories with different indices of refraction, which changed their relative speed of travel within the medium, altering the differential group delay element and linear displacement measured at the receiver location upon their return path from the loop transducer.

DESCRIPTION OF THE FIGURES

FIG. 1 a complete depiction of the present invention. The fiber sensor loop is shown with 10, encircling an electrical conductor shown with 12 which rests on an insulator support 13 at a location shown with 6, inside of a weather-proof flexibly armored jacket shown with 14. The fiber loop shown with 10, 14 has extending and rigid end-reinforcing connector sleeves, shown with 2, which rest on the sensor support stands shown with 4 and plug in to the recessed fiber optic sensor loop connection ports, shown with 3 which are shielded from electrical field influences with the detachable hollow shell insulator covers depicted with 18. The fiber loop comprised of 10, 14, 2 continues through the internal routing of the extending fiber loop support arm shown with 5, 7. The entire fiber loop support arm extension comprised of 4, 5, 7 is statically connected to the toroidal sensor base shown with 9, which mounts through the center 15 to the insulator bushing support column shown with 11 and is supported by the rigid and solid support region shown with 17, where 11 is supported by cross-arm mounting hardware shown with 8 on the crossarm 16. The toroidal sensor base 9 has internal routing around its hollow perimeter for the continuation of the fiber loop 10 to the auxiliary/external transmit and receive ports shown with 1 which terminate the polarization maintaining optical waveguides 20 which are routed internally within the device, starting from the optical connector ports 3. The TX/RX ports 1 are for external conduit-routed fiber connections from the SCADA monitoring center, and comprise a complete loop around the power conductor 12, and connect to a high speed fiber backbone link with bidirectional passive optical splitters, indexed to unique frequencies corresponding to different sensor locations. 21 shows a 90 degree linear light polarizer connected inline with the internally routed waveguides 20, which the transmitted unpolarized light pulses pass through after entering the TX/RX input 1 before travelling through the fiber transducer loop 10 around the power conductor 12 via the optical ports 3. 22 shows an optical beam splitter connected inline with the internally routed waveguides 20, at a location directly before the input stage of the linear polarizer 21, with a dual output from the beam splitter 22 connecting in parallel to the input of the linear polarizer 21 and a reference photon waveguide 24 which encircles the conduit toroid ring 9 only, and does not pass through the polarizer 21 or the transducer loop 10, and connects with an optical reference connection port 23, and creates an isolated and separate waveguide path from that used by the rotated polarized light which has travelled around the transducer loop 10.

FIG. 2 shows an alternative embodiment of the present invention, wherein each sensor base support stand 4 connects with an individual support arm extension 5, such that the toroidal sensor base 9 connects directly with two extending support arms 5.

FIG. 3 is a depiction of the present invention without the insulator covers 18, and shows the reinforced fiber loop ends 2 connecting with the optical ports 3 of the sensor stand 4.

FIG. 4 shows an alternative embodiment of the present invention, wherein each sensor base support stand 4 connects with an individual support arm extension 5, such that the toroidal sensor base 9 connects directly with two extending support arms 5 and is a depiction of the present invention without the insulator covers 18, and shows the reinforced fiber loop ends 2 connecting with the optical ports 3 of the sensor stand 4.

FIG. 5 is a depiction of the optical current monitoring system, based on wavelength division channel multiplexing and passive optical network architecture. The control center, shown at far left, transmits polarized light at multiple wavelengths within a transmission spectrum, across the horizontal backbone fiber link which connects to all poles shown, and comprises the horizontal communication link between all power pole current sensing locations and the control center. Passive bidirectional optical splitters are mounted on the poles at the box-locations shown, and optical wavelength filters allow each fiber loop sensor to conduct an optical wavelength unique to its sensor identity, and which is then transmitted back to the control center with a polarization angle rotation proportional to the magnitude of electric flux present on the live conductor at the sensor location.

FIG. 6 is a communication block diagram depiction of the metering process for deploying the sensor along a power line. Using the passive optical network topology with bidirectional optical signal splitters and wavelength attenuator filters on each pole, shown in FIG. 2, the utility control center transmits polarized light waves, with measured and known polarization angles and across a multiplexed wavelength spectrum, through the fiber loop sensors, which then is received back at the control center, where the difference between the transmitted and received optical polarization angle for each sensor wavelength is input to a microprocessor for electrical state estimation of current quantities within the sensor network.

FIG. 7 shows a 3-phase utility pole Fiber To The Transducer (FTTT) cabling configuration, where a typical pole will have a junction box with pass through optical couplers, splitters, and demux wavelength filter units, shown as rectangles, which tap a portion of the signal spectrum from the horizontal high-speed data link “transmit” fiber and couple it with a vertical fiber riser segment. This tapped and filtered signal is routed up the pole via the bidirectional BiDi fiber riser and upon reaching the primary crossarm the fiber splits into connectorized and pre-terminated patch-cord segments which plug in directly to the “TX/RX” input terminals of the present invention, where the polarized light travels through the internal optical conduits of the present invention along opposite paths, traverses the fiber transducer loop of the present invention along counter propagating paths, which encircles the flux path of the electrical phase conductor, travels back to the “TX/RX” output terminals of the present invention by its continuous internal optical routing, then re-couples with the single bidirectional BiDi fiber vertical riser return path via the connectorized patch cords and travels back down the pole and re-couples with the return fiber path of the main horizontal data link backbone of the sensor network through a BiDi bidirectional fiber transceiver which couples the two signals comprised of the counter-propagating polarized light waves into a single signal output, where the horizontal data-link is duplexed, with separate transmit and return fiber channels, to avoid signal interference, and where the transmit path will have an optical attenuator at its termination, where the linear sensor network ends, to eliminate the possibility of back-reflectance to the source laser.

FIG. 8 is a cross-sectional view of the toroidal sensor base 9 of the present invention and depicts the mounting configuration with respect to the insulator column 11 and crossarm 16, where the insulator support column 11 has a flanged support platform which the rigid structural region 17 is supported on while the hollow center 15 connects to 11 in a bushing style mechanism.

FIG. 9 is a profile view of the present invention, as viewed from a co-linear perspective with a monitored electrical conductor.

FIG. 10 is a cross section and profile view of the fiber transducer loop. 14 shows the flexible outer shielding, made from material such as outdoor-rated polyvinyl chloride (PVC), with embedded kevlar string. 25 shows the outer extents of a vibration-damping insulation layer, to minimize vibrational effects on the optical waveguide 10. 26 shows a loose buffer tube which would contain a water-blocking gel, encased within the flexible outer armor 14 and vibration-damping insulation 25.

DETAILED DESCRIPTION OF THE INVENTION

The center 15 of the sensor base 9 connects to the insulator support column 11 with a bushing mechanism. In practice this may require special insulator support columns fabricated with threads which 15 screws on to securely attach 9, or a flange support integrated with the base of the insulator support column 11, which supports the center-proximate mechanically rigid and solid region 17 of the center-distant hollow and toroidal sensor base 9.

The sensor base 9, 15 and the fiber sensor support extensions 4, 5, 7 are mounted to the insulator support column 8, 11. The fiber sensor loop 2, 10, 14 is connected to the rest of the device at the recessed, weatherproof connectorized attachment ports 3. After plugging in to 3, the fiber loop sensor 2, 10, 14 continues internally through the device, as 10 only, to the auxiliary signal transmit and receive ports 1, located on the sensor base 9.

The optical beam splitter, shown with 22, is connected inline with the internally routed optical waveguide 20, after the TX/RX SCADA input stage shown with 1, and housed and contained within the sensor base toroid conduit ring 9. The beam splitter has twin parallel outputs: one connects to the input stage of the linear optical polarizer shown with 21, another connects to a reference waveguide 24 which is routed within the sensor base conduit ring 9 and connects to an optical connection port 23 located on the exterior of the sensor base. The photon output from the beam splitter 22 which does not pass through the linear polarizer 21 and which does not travel around the fiber transducer 10 is a reference for comparison with a co-generated photon which does travel through the polarizer 21 and the fiber transducer 10, and the former unpolarized reference photon travels along a reference waveguide, shown with 24, to a separate reference photon outlet port, shown with 23, while the latter polarized and rotated photon travels through the linear polarizer, shown with 21, and around the fiber transducer loop, shown with 10, via the optical connection ports, shown with 3, and returns to an opposite TX/RX port, shown with 1, from the input feed to the sensor loop signal path, via the internally routed optical waveguide, shown with 20.

Data traffic on the horizontal backbone link, which connects the control center transmitters and receivers to the sensor loop network, is structured such that the bi-directional optical splitters which tap off to the individual fiber loop sensors at the pole location are the only potential sources of return signal traffic on the horizontal link to the control center receiver.

Each optical attenuator in series with the incoming signal feed to a fiber loop from the horizontal backbone filters every wavelength but one, which is unique for a sensor. This occurs before the polarized light test signal from the control center transmitter is routed around the conductor. A fiber sensor loop only conducts a single wavelength, which is transmitted at the sensor base as a return signal to the bi-directional optical splitter, which reflects and passively transmits the light wavelength which has passed around the power conductor back to the control center receiver, where the polarization rotation of the light can be measured and calculated with for electrical state estimation by microprocessor computers.

The control center transmits polarized light on a multiplexed channel across an indexed frequency spectrum, and that unique wavelength bands within this spectrum can be assigned to different sensors within a network. This multiplexed spectrum of polarized light is transmitted across a horizontal optical signal link which connects all utility poles within a network.

Bi-directional optical splitters tap off the horizontal link at a pole sensor location and transmit the signal through an optical attenuator which filters all wavelengths except for the channel band assigned to the sensor at the SCADA address of the pole sensor location. Bi-directional passive optical splitters along the horizontal link are the only sources of return data traffic to the control center receiver.

By filtering the incoming received sensor signal, which a bi-directional optical splitter taps from the long haul horizontal backbone link, with an optical attenuator which only transmits a wavelength particular to a unique sensor, the entire transmitted spectrum is returned to the control center receiver, but with only one signal per data channel.

Because any wavelength is theoretically attenuated at all locations along the passive optical sensor network except at the location of the sensor assigned to it, the data integrity of the returned signal is preserved across the transmitted channel spectrum.

All Components of the Device are Fabricated with a Polymer Material Having an Electrical Insulation Rating Exceeding the System Voltage of the Device Application

Each pole which is current monitored has a fiber junction box with pass-through optical couplers, which tap a portion of the light signal transmitted across the high-speed data link backbone of the metering network. An optical filter selects for the wavelength channel band which has been addressed and assigned to the pole in question. Bend-insensitive single mode fiber is then routed vertically, from the pole fiber junction box, up to the primary cross-arm where the three conductor phases, and optionally a neutral, are supported by pin insulators, at the base of which the toroidal base of the present invention is attached. At the primary cross-arm level, the single-mode fiber, which is transmitting polarized light, splits into 3 or 4 connectorized terminations, representing a signal power division at this junction of ⅓ or ¼, in dBm, which enter the “RX” input of the present invention, traverse its transducer loop path, and exit the “TX” output as an individual bend-insensitive single mode fiber strand, and the 3 or 4 individual transducer phase “TX” outputs converge on the primary cross-arm, at the same location where the fiber phase inputs split, and a single bend-insensitive fiber carries the polarized light pulses from all 3 phases, and optionally a metered neutral, down the pole to the fiber junction box, where an optical coupler directs this light into the return path of the high-speed datalink backbone, returning to the SCADA receiver and control center where metering calculations are performed.

There is a potential for a large number of mechanical connections in the network described, as the transducer itself contains 4 connector points where signal loss occurs: 2 at the plug-in connections of the transducer loop to the device's support platforms, and 2 at the TX/RX terminals on the toroidal base. The optical couplers in the fiber junction boxes will cause signal attenuation and power loss, and the splitting of the single-pole signal into the individual phase components reduces the incident signal power, in dBm, by a factor of 3 at the point of individual phase metering, or 4, if the neutral wire is being metered. For this reason, the power budget of the overall system must consider all connection loss points, and the power rating of the laser transmitter will provide for a minimum level of light transmission across each transducer such that the returned signal to the SCADA monitoring computer is detectable.

In a 3-phase alternating current distribution network, under normal balanced load conditions with no faults occurring, the voltage and current magnitudes are all equal, represented as either rotating phasor vectors or oscillating sinusoids. These equal magnitude current and voltage vectors are displaced equally by 120°, and phase rotation can be either “A-B-C” or “C-B-A”, which is either clockwise or counter-clockwise in the phasor domain. Viewed as sinusoids, the leading phase peaks first, on the horizontal time axis, and the lagging phases peak later, or afterward, on the time axis. The transducer device passes a stream of polarized light pulses around the magnetic flux vectors which are generated by the electric field, which exists due to the voltage potential applied to the phase wire by its generation source, which causes a circular rotation of the polarized light pulses, or a change in their polarization angle. Assuming that this rotated pulse of polarized light can be transmitted without undue delay back to the SCADA receiver, it now contains information about the magnitude of magnetic flux in the electrical phase conductor at the moment in time when the light pulse traversed the transducer fiber loop, based on the Faraday rotation effect. Then each pulse of light can be analogously compared to a digital sample of the analog current signal, which represents the electrical power and loading present on the phase conductors, after correlating the degree of measured polarized light rotation with an inferred magnetic flux density value, using Faraday's equations relating the optical and magnetic quantities. Assuming that the polarized light splits evenly among the 3 or 4 “RX” inputs on the transducer, and, critically, re-couples into the single bend-insensitive fiber riser which is the pole's vertical return signal conduit, without wave-mixing, super-position, interference, reflection, or excessive disruption to the time-domain ordering of the pulses, then all 3 phases can be sampled at once, while distinguishing phases, because they are phase displaced in the time domain! For a 10 Mbit/sec sensor network speed, this equates to a sampling rate of 10 million pulses for second. Considering that the phases are only 60 Hz at the fundamental frequency, this provides a theoretical sampling rate of 16,667 transduced light pulses per wave-cycle, and perhaps can provide an operating margin for a non-zero bit error rate, as there are an abundance of individual time-based data points for any given wave cycle. Assuming the polarized light from the transducer output of all 3 phases can be coupled back into the pole's single-mode fiber return path and transmitted to the SCADA receiver via the optocoupler connection in the pole's fiber junction box which connects with the high speed sensor network horizontal data link, then, as a broad generalization, the map or graph of the phase current signals which are inferred from the polarization angle shift of the rotated polarized light pulses, would be a combination of high, low, and zero states, corresponding to the sinusoidal peaks, troughs, and zero axis crossings of the sinusoids, and because the sampled phase current signals are displaced equally by 120 degrees, there is no superposition of the transduced polarized light signal outputs, as each phase has a different magnetic flux state at a given point in time, resulting in unique and differentiable polarization angles for the returned polarized light pulses, which occur and exist at different magnitude, or Y-axis, points on a time-domain plot of the sinusoidal current phases, such that over millions of samples, the 3 phase sinusoids become distinguishable and differentiable. This assumes that there is no undue delay in the light signals returning to the SCADA center, and that all 3 phase's contemporaneous transducer outputs arrive synchronously at the SCADA receiver. Where each pole taps a portion of the main data-link light signal spectrum, filters and selects for the wavelength channel-band addressed to the pole, the signal power must split equally at the primary crossarm among the patch cord transducer input cables, from the single-mode fiber vertical riser, and then recouple into the vertical riser from the transducer output patch cords, without superimposing, wave-mixing, disordering, or back-reflecting, to preserve the sampled time-domain signal integrity of the 3 phases. If these conditions are met, then millions of light pulses per second will map and illuminate the sinusoids as separately identifiable signals, by nature of their displaced, non-superimposed nature.

A practical consideration inherent with the linear point-to-point nature of the horizontal passive optical sensor network is that poles which are more distant from the SCADA transmitter laser and receiver will have a natural delay in their signal return time, while poles which are closer will return signals faster. This can be compensated for in the SCADA calculations, based on the known distance of each pole metering location from the SCADA transmitter and receiver, using the average speed of light for the wavelength channel assigned to the pole and its metric linear distance, to infer how far back in time the received light pulse traversed the phase magnetic flux path, and the true time-domain point in the phase current sinusoid the pulse represents, via its altered polarization angle correlated with magnetic flux density and electron flux in terms of charge migration rates.

To prevent the individual phase sensor light pulse outputs from interfering, superimposing, or back-reflecting on their return path down the vertical fiber riser, when traveling from the primary cross-arm patch cord breakout and junction point, ribbon fiber which contains multiple individual fiber strands shall be used for the vertical fiber riser return link, which transmits the rotated polarized light pulses from the sensor output, which are in the wavelength channel band which was filtered for the sensor location wavelength address, back to the horizontal data-link return cable, which directs photon traffic to the SCADA receiver, such that each individual sensor output has a dedicated fiber strand channel for its coupling into the horizontal backbone which interconnects all sensors in the passive network with the main SCADA laser transmitter and photodetector receiver.

Multi-fiber opto-couplers are required to connect the sensor output patch cords and associated multi-fiber vertical fiber riser return link with the horizontal backbone data-link cable in the pole fiber junction box, such that each phase transducer light pulse output couples into the multiplexed horizontal backbone through an individual fiber strand, to preserve signal integrity and avoid excessive bit error rates at the SCADA receiver. To protect the vertical riser forward-to-the-sensor and return-to-the-horizontal-backbone data fibers from damage, along with all individual phase sensor breakout patch cords, all cabling shall be of the loose tube, gel-filled water blocking, and flexibly armored variety, with PVC or similar jackets, to ensure long term durability of the cable when facing animal or environmental threats. Four-strand armored breakout cable with water-blocking and a pre-installed sensor patch cord break out splitter for the primary cross-arm sensor patch-cord junction point could be fabricated and used alternatively, for the vertical riser sensor output return data link, and cabling designs for routing individual fiber strands from the sensor output to the horizontal data-link via a multi-fiber optical coupler in the pole's fiber junction panel will be obvious to one of ordinary skill in the art field of the present invention, given the aforementioned environmental protection and signal-routing requirements.

The fiber optic waveguide type used for the forward and return paths of the horizontal data-link backbone, and for the vertical riser links at the individual pole sensor locations, shall be single-mode and of the Polarization-Maintaining variety, where such Polarization-Maintaining fiber preserves the polarization state of orthogonally polarized light modes and prevents pulse mode spreading. The type of fiber used for the transducer loop which encircles the electrical conductor and plugs in to the base of the sensor shall be single mode and Bend-Insensitive (BI), where an optical trench prevents light modes from exiting the cladding due to a macro-bend in the fiber. The transducer loop is not Polarization Maintaining, as its polarized modes are intended to rotate and experience a relational displacement in the presence of the magnetic flux which is proportional to the conductor current. If macro-bends and mechanical stresses are minimized within the fiber sensor network, then the transducer loop is the only location where significant light mode polarization can occur, which provides measurement certainty and reduces error sources in the signal path.

All plasticine device components for the transducer loop and sensor shall be constructed from polymer insulator materials with a dielectric strength sufficient to remain a strong insulator at the system voltage level of the component application. No metallic components may be present. Precision ceramic ferrules may be used for fiber alignment at the reinforced connector end-points of the transducer loop which plug in to the sensor base, and at all other fiber termination connector points on the sensor. In the presence of high voltage, plastic polymers normally used in fiber optic hardware fabrication will experience dielectric break-down and be mechanically compromised, thus fabricating the connector hardware and sensor receptables from the polymer material types used for high voltage insulator disks is a construction requirement, though this will be obvious to one of ordinary skill in the art field of the present invention.

The passive optical wavelength channel filters and opto-couplers described are a mechanical solution for signal MUX/DEMUX operations, which are required to tap and then re-couple the wavelength channels which are used to transduce electric current at individual sensor locations, with respect to the transmitted and received, or forward and return, paths of the horizontal SCADA data-link spectrum. A MUX and DEMUX passive optical switch, capable of multiplexing a single received polarized light signal of a specific wavelength channel with an entire signal spectrum containing polarized light signals of multiple channels, such as when recoupling the transduced sensor light modes with the return path of the SCADA horizontal data link, or demultiplexing one polarized light signal within a specific wavelength channel at a time from the forward path of the SCADA horizontal data-link signal spectrum, such as when band-pass filter selection for the wavelength channel assigned to a sensor location occurs, prior to current transducing, would be ideal for this application, in order to prevent wave-mixing due to light mode superposition at the coupling and decoupling points at a utility pole fiber junction box within the sensor network.

To protect the reinforced fiber transducer loop ends from stray electric field influences, and prevent signal noise injection after the transduced light pulse has completely traversed an entire loop around the electric conductor and transduced the electric current magnitude into a proportionate photon signal, based on the degree of axial rotation induced between the two polarized light waves, relative to their respective planes, hollow insulator covers are attached to the sensor support stands after the transducer ends are plugged in to the recessed optical connection ports of the sensor support stands, and shield the entire exposed surface area of the support stand from the electric field of the energized electric conductor. The detachable hollow shell insulator covers are also weatherproof to provide an additional layer of water-blocking protection for the recessed optical connection ports and the reinforced fiber transducer end junction point. Additionally, the shape of the insulator disks will provide an aerodynamic profile which produces less drag force due to air molecule fluid friction in high wind events, based on a velocity profile which is more likely to be laminar and less susceptible to fluid turbulence.

The common mode differential phase shift measuring scheme comprised of iso-rotational and counter-propagating circularly polarized light waves requires bidirectional (BiDi) single wavelength fiber links to transmit data to and from the pole mounted sensors, and single wavelength BiDi transceivers which split or couple the output signal based on a sensed ingress or egress wave property, based on the forward or reverse direction of the travelling wave relative to the transceiver input, such that the tapped and filtered circularly polarized light signal from the horizontal SCADA link forward path is split into two separate outputs, which feed in parallel to the “TX/RX” signal contacts and connection points of the claimed invention. On the return path, the bidirectional BiDi fiber waveguides of the transducer loop and internally routed optical waveguides of the claimed invention, and the return link along on the fiber riser, are re-coupled from dual signal inputs into a single signal output, by another BiDi single wavelength fiber transceiver, and this combined signal output which contains the data for the phase displacement measured for a specific time and pole location is coupled with the return path of the horizontal SCADA data link and received at the central monitoring point for current calculation.

A simpler alternative to the dense wavelength division multiplexing scheme discussed, which requires optical splitters and filters to perform the mux and demux operations, and calculation-based compensation for the wavelength-dependency of the Verdet constant of the transducer loop of the present invention, would be to route a single bidirectional fiber to each sensor, within a shared aerial conduit assembly. The advantage of this as compared to regular signal or telephone wire is the long-distance range of optical signals, which still enable a passive sensor network, whereas conventional electronic signals would require signal repeaters and separate power sources, and preclude passive network architecture. The ability to use pure fiber optical cables to connect to the primary voltage sensor base of the present invention is an additional advantage not possible with electronic signals and metallic conductors. As the present invention is constructed from polymer materials with an insulation rating greater than the system voltage, the internal optical waveguides are shielded from stray electric field effects which could rotate the polarization vectors of the light waves and introduce noise into the transduced signal, which also enables an all-fiber optical sensing network to extend to the primary voltage level without induction hazards and the risk of arcing or equipment failures, as there are no metallic components present in the device or fiber riser cable shields which connect to the data ports of the present invention.

The device may require avian deterrence in practice, though the need and best practice for achieving this will be obvious to one skilled in the art field of the present invention.

Assume a continuous function, which maps the polarization angle between two linearly polarized light modes, to the measured differential group delay element (DGD) between said linearly-polarized modes, which is based on a known and continuously variable index of refraction within the waveguide medium, due to light mode linear polarization angle, from waveguide material birefringence within an optical fiber, where the index of refraction varies as a continuous function of linear polarization angle.

Two orthogonally polarized light modes, transmitted across polarization maintaining fiber, will arrive at a forward point at a theoretically assumed time, and with a calculated differential group delay element, based on the polarization-angle-dependent variable indices of refraction of the transmitting medium, and the linear distance to the forward point in question.

Considering a return path, from said forward point, to the original transmitting location of the orthogonally polarized light mode, across polarization maintaining fiber, which is theoretically immune to material stress induced birefringence: the differential group delay element, as measured for the returned linearly polarized light pulse, is an indicator of polarization-angle change, at the forward point location in question. Assuming that the index of refraction is mapped continually, throughout a waveguide medium, as a function of linear polarization angle, the relative angle of polarization, between linearly polarized light modes, can be inferentially calculated, based on the differential group delay element measured between the two modes.

The difference in differential group delay element, between two linearly polarized light modes, as observed from an origination location, between two transmitted linearly polarized light modes, and received light modes, upon return from a forward point in question, is thus a theoretical indicator of the relative change in polarization angles, between the two linearly polarized light modes, occurring at the forward point turnaround location in question.

The differential group delay element, between two linearly polarized light modes, across a polarization maintaining waveguide medium, is a theoretically assumed and calculated quantity, and is a function of known material birefringence variation as a function of polarization angle. For a linearly polarized light pulse returning to an original transmission location, within a polarization-maintaining fiber medium, the measured differential group delay element of the received polarized light pulse, from its return path, provides transduced data regarding the relative change in polarization angle between the two linearly polarized light modes.

$\begin{matrix} {n = \frac{1}{\sqrt{\frac{\cos^{2}\theta}{n_{0}^{2}} + \frac{\sin^{2}\theta}{n_{e}^{2}}}}} & {{Eq}.\mspace{14mu} 4} \end{matrix}$

Where:

-   -   θ=polarization angle         -   n₀=ordinary idex of refraction,         -   associated with unpolarized light, travelling along the             ordinary optical axis, which is the zero angle reference for             the polarization angle coordinate axes.     -   n_(e)=extraordinary index of re fraction, associated with the         extraordinary polarized axis which is rotated at angle θ from         the ordinary optical axis, as represented with vector notation.

The differential group delay element is a time or distance quantity. Only polarized light modes travelling along the extraordinary axis will rotated in the presence of an electromagnetic field, relative to the ordinary optical axis zero reference. The light mode travelling along the ordinary axis will not rotate. The change in relative angle between the linearly polarized light modes which are travelling along the ordinary and extraordinary axes is induced by an electromagnetic field. Light can be polarized linearly at the input stage with a known angle, such as 90 degrees. The polarized light mode travelling on the extraordinary axis will rotate proportional to the magnitude of the magnetic field, as described by Eq. 1. To measure the degree of rotation, relative to the arbitrary input reference value of 90 degrees, the observed differential group delay at the receiver location is used: the unpolarized light component travelling along the ordinary optical axis arrives at an expected and calculated value, based on n₀=n for unpolarized light, and is a material property with known values. When the receiver detects light pulses at time points or intervals which are not consistent with the digital frequency pattern expected for a given value of n and the bit-rate, these are assumed to be the light pulses which are travelling along the extraordinary axis, and which are polarized. To find the polar rotation angle θ of the extraordinary axis, the index of refraction n_(e) is used, and n_(e) is found from the differential group delay element, Δτ, for the polarized light modes, which is the difference in arrival time between the rotated pairs.

From a given transmitter location, to a given sensor location, an unpolarized light pulse travelling along the ordinary axis with rotation=0 will traverse the distance between said location according to

$\begin{matrix} {t_{0} = \frac{dn_{0}}{c}} & {{Eq}.\mspace{14mu} 5} \end{matrix}$

where d=distance between transmitter and sensor, n is the normal index of refraction for the fiber, along the ordinary axis and with zero polar rotation, and c is the speed of light, 3e8 m/s. To calculate n_(effective) a value of t is used in Eq. 5 which is the sum of the time value calculated based on n₀ and the measured differential delay element time value, which is the phase shift between the two wave numbers of the polarized modes, while d and c are unchanged, the calculated index of refraction n_(effective), where:

$\begin{matrix} {t_{effective} = {t_{0} + {\Delta\tau}}} & {{Eq}.\mspace{14mu} 6} \\ {\frac{t_{effective}c}{d} = n_{effective}} & {{Eq}.\mspace{14mu} 7} \end{matrix}$

The differential group delay element is seen as two distinct bit frequency patterns, as for linearly polarized light, the components travelling along the ordinary and extraordinary will arrive a fixed forward location at different times, from material birefringence and different indices of refraction and resulting wave propagation velocities within the fiber medium. The phase-shift between the two digital pulse signals, as a time value, is the observed differential delay element magnitude. The polarization angle change Δθ=90−θ from Eq. 3. The current I is then found with Δθ in Eq. 2 and Eq. 3.

While the value of n used in Eq. 4 is calculated using Eq. 5, Eq.6 & Eq. 7, values of n_(e) would be experimentally determined and measured parameters for a given optical material, and swept for all values of θ, such that distinct value-pairs are mapped for all {θ, n_(e)}, and Eq. 4 can be solved iteratively to estimate the value of 0 corresponding to the effective refractive index n calculated with Eq. 5, 6 & 7.

Alternatively, the polarization angle θ of the rotated light after it travels through the fiber transducer loop of the present device can be measured directly with a polarization angle meter, and existing instruments in the art field of the present invention can perform this measurement function and will be obvious to one of ordinary skill in the art field of the present invention.

For purposes of the previously referenced time-distance birefringent wave-delay calculations, it is desirable to have a reference photon for measurement comparisons, which originates at the location of sensor measurement, contemporaneous with the polarization of the transduced and rotated light mode produced at the sensor output.

In the preferred embodiment of the present invention, an optical splitting stage directly precedes the input of the linear polarizer, and occurs after the TX-RX input stage present on the toroid conduit ring device exterior, with an output connected to a separate optical waveguide medium which is housed within the toroid conduit ring, with a path not including the fiber transducer loop of the present invention, and remaining unpolarized, such that an unpolarized photon pair exists for each linearly polarized and transduced photon.

The unpolarized photon, which travels on a waveguide routed around and within the toroid conduit ring, connects to a reference output, for co-transmission with a linearly polarized photon twin from the fiber transducer output.

For the case of the preferred embodiment of claims 1, 3 & 4, where the outer toroid conduit ring of the present invention houses and contains a beam splitter connected inline to the TX-RX external input from the SCADA unpolarized light source, with parallel outputs from the beam splitter connected to a linear optical polarizer and to a separate all fiber waveguide which links to a separate output terminal on the ring conduit exterior of the device, and the output from the linear polarizer is routed through the fiber transducer, and back to a separate TX-RX sensor output terminal: the unpolarized photon within the pair, which is generated after the beam splitter and transmitted along the separate fiber waveguide to an optical outlet terminal located on the device exterior, can be routed within and around the toroid conduit ring a distance exactly equal to the path-length of the polarized photon which traverses the fiber transducer loop, such that there is no path length imbalance resulting in a phase delay in arrival time between the polarized-rotated and unpolarized-reference photon pairs. Alternatively a return path length imbalance from the pair-generation location of the beam splitter located within the sensor toroid housing can be measured and compensated for in calculations.

The purpose of Eq. 1 to Eq. 7 is to infer the electrical current flowing in a live conductor, based on measurement data from an all fiber single mode loop transducer, of the polarization angle rotation change of light passing through said transducer, which is attributable and proportional to the magnetic field flux density which surrounds the energized conductor, as observed at a known distance from the conductor surface.

The unpolarized photons are generated at the sensor location, and are a fixed location reference for telemetry calculations, as they travel along the ordinary optical axis with a known and constant index of refraction, and will travel across a fiber link of known distance with constant velocity.

The polarized photons which are generated by the linear 90 degree polarizer which is connected inline with one of the parallel dual outputs of the sensor beam splitter will traverse the fiber transducer loop and experience a rotation angle change relative to the 90 degree reference input. The linearly polarized photon output of the fiber transducer loop will travel at a different velocity than an unpolarized photon along a birefringent fiber medium, and the difference in velocity between the unpolarized reference photon and the polar-rotated and transduced photon, within a given pair, can be used to infer the difference in refractive indices as a function of extraordinary optical axis, which with Eq. 4 depends on the optical polarization angle θ, which is the primary measurement variable of interest.

The creation of a reference photon to pair with the transduced signaling photon is the basis for common mode sensing, and noise cancellation is possible by measuring dispersion or rotation seen by the unpolarized reference photon and subtracting these signals from the background of the polarized and rotated photon pair.

The output of the sensor, as seen at a TX/RX optical connection port 1 which connects to the internal waveguide end which is the exit point for photons which have travelled around the fiber transducer loop after passing through the linear polarizer, provides linearly polarized light which has travelled a loop path around a magnetic field of significant flux density. The Verdet constant of an all fiber waveguide transducer can be manipulated with the addition of dopants, and assuming a transducer with sufficiently large Verdet constant, the polarized light transmitted to the output of the sensor base contains a direct measurement of θ for calculations with Eq. 1, 2 & 3. Measuring the polarization angle change relative to the 90 degree reference input, Δθ, directly from this signal output stage is the overall usage intention of the preferred embodiment of the present invention, and preserving the signal integrity after the sensor output stage, and ensuring noise immunity during transmission over distance, are design implementation challenges which are outside the scope of the claimed present invention.

For linear polarizations, the angle θ expresses the angular displacement between the ordinary and extraordinary optical axes, which the polarized light modes travel along. A mode travelling along the ordinary axis experiences no angular rotation, or displacement about a reference point, in the presence of an electric or magnetic field, while a mode travelling along the extraordinary axis does, such that the relative angle between the linearly polarized modes travelling along the stationary, or ordinary, and rotating, or extraordinary, optical axes will shift, and when this occurs in the presence of a charged conductor it is the basis for current transducing using Eq 1, 2 & 3. From Eq. 4, the effective index of refraction for polarized modes is a function of the polarization angle, or the angle between the ordinary, or reference, and extraordinary, or measurement, axes. To infer a change in polarization angle, relative to a known reference value, of a linearly polarized photon, it is only necessary to observe its velocity difference relative to an ordinary optical axis standard, in order to calculate the polarization angle, θ, as a function of the extraordinary axis angular position, and the polarization-angle dependent index of refraction, based on a known waveguide birefringence profile.

To measure polarization angle using differential wave propagation velocities, a reference cable of sufficient length to allow linear separation to occur between the ordinary and extraordinary modes, as a function of their different experienced indices of refraction, can be used, where the length requirement of the reference cable is determined by the time-resolution measurement capabilities of the photodetector.

The birefringence property exploited by said measurement system is based on material anisotropy within the glass waveguide medium, where the grain-boundary between silica atoms is not uniform spatially, and interstitial atomic defects, or dopants, interact with a forward propagating wave to alter its trajectory and velocity, based on nano-scale collisions between the sinusoidally propagating photon particle and the defects in the silica crystal grain boundaries which the wave passes through. A fiber transducer would be calibrated such that a correlation is measured between the effective index of refraction, and the angle of polarization between the ordinary and extraordinary linearly polarized light components, for the entire range of light polarization angular displacement within the waveguide. 

1: A device which installs a passive fiber optic current sensor on a utility pole crossarm insulator pin, below and in auxiliary configuration with, a power line insulator, and which is fabricated entirely from a ceramic or polymer insulating and non-conductive material, comprising: A sensor base, featuring: A hollow center location, of a polygon shape which is geometrically congruent with an insulator pin hardware base, A solid and rigid structural support plane, which connects with and extends radially from, said center location, A toroidal conduit ring, which integrates at an inner circumference location with the structural support plane at an outer circumference and perimeter of said support plane, which has a plurality of optical connection ports integrated at an accessible location on the exterior of said conduit ring, and where said optical connection ports terminate an internally-routed optical circuit, A hollow cylindrical support column, which concentrically surrounds the insulator pin hardware base to form a contact surface with a top region of a utility pole crossarm and which creates a support base for the entire device; An optical fiber transducer cable assembly, featuring: A waterproof and armored outer cable jacket, An inner layer of vibration damping material with thermal insulating properties, A bend insensitive single mode optical waveguide with a non-zero Verdet constant, encased within said jacket and insulation, A pair of transducer cable ends, with rigid material reinforcement attachments and optical port connectors, where said connectors terminate the optical waveguide; A pair of transducer support platforms, featuring: An optical connection port for each end of the transducer cable assembly, An attachment mechanism for a covering surface, where said covering surface can shield the transducer cable assembly ends from electromagnetic interference and gas or liquid infiltration; and An extending rigid support conduit, featuring: A routing path for the internal optical circuit, which is compliant with a minimum bending radius of an optical waveguide, An end which integrates with the toroid conduit ring, An opposite end which branches to form a pair of connections with the transducer support platforms, at a height such that the optical connection ports located on the platforms are displaced below a power line conductor center by a distance equal to the radius of a complete loop formed by the transducer cable assembly, when said transducer encircles an energized power line conductor, with a connection between the conduit and the transducer support platform having a structural geometry which is compliant with a minimum bending radius of an optical waveguide. 2: The device of claim 1, wherein the branching support conduits, which extend toward the conductor and connect with the fiber transducer loop support stands, connect directly with the outer toroidal base, such that the outer toroid of the sensor base has two support extensions directly connected to its structure. 3: The device of claim 1, wherein a linear optical polarizer is connected inline with the internal optical waveguides, and housed within the toroidal conduit ring, and at a light path location before the fiber transducer loop. 4: The device of claims 1 and 3, wherein an optical beam splitter directly precedes an input stage of the linear optical polarizer, and said beam splitter has an output which connects directly to an optical waveguide, while an opposite end of said waveguide encircles the outer toroid ring conduit, and said device has an additional recessed optical connection port integrated with the exterior of the outer toroid conduit ring, which connects with the opposite end of said waveguide and directly links an output stage of said optical splitter with said third optical connection port. 